Dynamic attitude measurement method and apparatus

ABSTRACT

A method and system senses the attitude of an accelerating object by measuring acceleration with accelerometers in three orthogonal axes and measuring angular rate with angular rate sensors disposed about each such axis to compute attitude of the object accurately relative to a vertical axis. A processor updates a quaternion representation of attitude based upon the angular rate of the object, and a corrective rate signal is determined from level frame acceleration as a reference for a Kalman filter in calculating the attitude of the object. When velocity or airspeed is available from an external source, an aiding algorithm is employed to provide accurate attitude representations throughout all flight regimes.

RELATED APPLICATIONS

This application is a continuation of application Ser. No. 11/026,256 (now U.S. Pat. No. 7,216,055) entitled “DYNAMIC ATTITUDE MEASUREMENT METHOD AND APPARATUS” filed Dec. 30, 2004 by Michael Horton et al. which is a continuation-in-part of application Ser. No. 10/684,950 (now U.S. Pat. No. 6,853,947) filed Oct. 13, 2003 by Michael Horton et al. which is a continuation of application Ser. No. 10/136,955 (now U.S. Pat. No. 6,647,352), entitled “DYNAMIC ATTITUDE MEASUREMENT METHOD AND APPARATUS”, filed on May 1, 2002 by Michael Horton et. al, which application is a continuation-in-part of application Ser. No. 09/326,738 (now U.S. Pat. No. 6,421,622), entitled “DYNAMIC ATTITUDE MEASUREMENT SENSOR AND METHOD”, filed on Jun. 4, 1999 by M. Horton, et al., which claims priority from U.S. Provisional Application Ser. No. 60/088,160, filed on Jun. 5, 1998, by Michael A. Horton, entitled “DYNAMIC ATTITUDE MEASUREMENT SENSOR AND METHOD”, which applications are fully incorporated herein by reference.

FIELD OF THE INVENTION

This invention relates to the measurement of attitude of accelerating bodies, and more particularly to attitude sensors and control systems.

BACKGROUND OF THE INVENTION

Certain known techniques for measuring and controlling attitude of a moving body commonly rely upon a gyroscope spinning about a vertical axis, or upon a liquid sensor, or upon a pendulum device responsive to downward gravitational orientation. However, the mass of a pendulum renders such devices also responsive to acceleration, and hence are not useful as attitude sensors in dynamic systems involving an accelerating body. Similarly, liquid sensors exhibit mass that affects attitude detection during acceleration, and also such sensors are vulnerable to vibration that affects surface characteristics of the liquid upon which sensing may depend.

Vertically-oriented spinning gyroscopes commonly operate as attitude sensors, but are usually heavy, bulky, expensive devices that are subject to precession and drift errors. They also suffer from poor reliability in rugged operating environments due to the moving parts that make up the technology which require periodic maintenance to keep the units operational.

Other known attitude sensors rely upon multiple GPS receivers at spaced locations to compute attitude from signals received at each location. However, such computation of attitude is subject to the distance inaccuracy of signals received at each location, and the spacing of the locations should be very much larger than the distance error associated with each such location, and this contributes to unacceptably large systems for making fine attitude measurements. Rate sensors of negligible mass such as ring laser gyroscopes have been used in attitude-sensing measurements, but are vulnerable to drift and associated long-term instability.

SUMMARY OF THE INVENTION

In accordance with the present invention, accurate attitude sensing is accomplished by measuring acceleration in three orthogonal axes and measuring angular rate about each such axis to compute attitude accurately relative to a vertical axis. Solid-state accelerometers and rate sensors are temperature compensated and are assembled into a small common housing for applications in rugged environments. Measurement errors attributable to fabrication misalignments, and the like, are calibrated out following initial assembly for highly reliable and accurate outputs from a compact, rugged assembly of components. Vibrating ceramic plates operate as rate sensors responsive to Coriolis forces to produce angular rate outputs independently of acceleration, and micromachined silicon devices operating as differential capacitors to sense acceleration in aligned directions independently of angular rate about the orthogonal axes.

A method in accordance with the present invention includes converting analog outputs of all sensors to digital values with stored calibration correction values. The signals representing total angular rate or rotational velocity about each of the orthogonal axes is integrated into a quaternion (i.e., a 4-element vector that completely describes the orientation of an object), and total angular rate is computed from the sensed and corrected rates. The direction cosines are computed from the quaternion, and the accelerations of the assembly are computed from the three acceleration signals multiplied by the direction cosines. Attitude and other parameters or orientation and motion of the assembly are derived from the data produced by the accelerometers and rate sensors within the common assembly.

In one embodiment of the present invention, a relatively inexpensive and compact-sized system generates an accurate representation of an attitude of an object. In particular, the system measures attitude for an object that may be accelerating, thereby overcoming the drawbacks of conventional attitude measuring devices mentioned above. Furthermore, such embodiment of the present invention provides a self-tuning system that automatically compensates for drift and that automatically updates the quaternion obtained from sensor outputs. The system generates highly accurate output data based upon measurements obtained from commercially available, low or mid-level performance sensors. In addition, the user of the system can provide input commands that can adjust the output data of the system in order to further compensate for factors in the environment of the system. This embodiment of the present invention also reduces the manufacturing complexity of attitude measurement devices by providing a calibration sequence that reduces the number of testing steps during the manufacturing process.

In another embodiment of the present invention, improved algorithms for attitude and heading calculations are based upon extended Kalman filter trajectory corrections, with accelerometers providing attitude reference information, and the Kalman filter providing corrections to the attitude trajectory as calculated from integration of rate sensor information. Extended Kalman filter algorithm involves intense calculations performed by a dedicated processor. A master processor calculates the attitude trajectory, and a dedicated or slave processor calculates the Kalman filter corrections and estimates of sensor bias. Resultant attitude errors are less than 0.1 degree under static conditions, and are a function of the dynamic acceleration profile under dynamic conditions. Typical results obtained under flight test conditions analogous to light-aerobatic maneuvers indicated only about 1-2 degrees RMS attitude errors.

DESCRIPTION OF THE DRAWINGS

FIG. 1 is a graph illustrating coordinate axes with respect to which the present invention responds to movements and orientations;

FIG. 2 is a block schematic diagram of one embodiment of the present invention;

FIG. 3 is a flow chart of an operational sequence according to the present invention;

FIG. 4A is a schematic diagram of one embodiment of the present invention for enhancing bandwidth;

FIG. 4B is a graph showing bandwidth compensation according to the present invention; and

FIG. 5A is a graph illustrating error correction over time under proportional gain control;

FIG. 5B is a graph illustrating error correction over time under fixed rate gain control according to the present invention;

FIG. 6 is a flowchart describing a method for determining the calibration coefficients and correction factors thereby providing a “factory calibration” used in accordance with the present invention;

FIG. 7 is a flowchart illustrating additional details of the quaternion update and normalization;

FIG. 8 is a schematic diagram of a system including co-processors for computing attitude trajectory and Kalman filter corrections;

FIG. 9 is a block schematic diagram of progressive stages of compensation of data suitable for extended Kalman filter processing;

FIG. 10 is a graph showing the vectors involved in calculating attitude error corrections associated with the body frame of a vehicle in relation to a tangent frame or local level horizontal frame;

FIG. 11 is a flow chart illustrating one component of an attitude error decision model according to the present invention; and

FIG. 12 is a flow chart illustrating another component of an attitude error decision model.

DETAILED DESCRIPTION OF THE INVENTION

Referring now to the graph of FIG. 1, there is shown a coordinate set of axes X, Y, and Z that designate directions of movement or orientations with respect to the ‘horizon’ 8 as a reference plane, and about which rotational motions are specifically legend as ‘pitch’ (i.e., rotation about Y in the XZ plane), and ‘roll’ (i.e., rotation about X in the YZ plane), and ‘yaw’ (i.e., rotation about Z in the X Y plane, also referenced as ‘heading’ or ‘azimuth’).

In accordance with the present invention, as illustrated in the block diagram of FIG. 2, solid-state accelerometers 9, 10, 11 are disposed in alignment with each of the X, Y, and Z axes, respectively, and inertial elements 13, 14, 15 are disposed to sense rate of change of angular displacement about each of the X, Y, and Z axes, respectively. The accelerometers 9-11 may each comprise conventional micro-machined silicon devices that operate on differential capacitance to produce an analog output indication of axial acceleration. Suitable devices are commercially available as Model No. ADXL05 from Analog Devices, Inc. of Norwood, Mass. Similarly, the inertial elements 13-15 are solid-state devices that each comprises a vibrating ceramic plate responsive to Coriolis force to produce an analog output indication of angular rate independent of acceleration. Suitable devices are commercially available as Model No. ENV-05H-2 from Murata Manufacturing Co., Ltd. in Japan. The accelerometers and rate sensors and a temperature sensor 17 may be assembled within a confining housing of about 3 cubic inches, or less, for unobtrusive installation in numerous applications. Optional magnetic sensors 18 a-18 c may be aligned with each of the X, Y, and Z axes in order to provide correction factors for heading (yaw), as described below. The analog outputs from the accelerometers 9-11, and from the inertial elements 13-15, and from the temperature-sensing element 17, and from magnetic sensors 18 a-18 c, are supplied as outputs 19 of the assembly, and are also supplied to an on-board Analog-to-Digital (A/D) converter 21 for conversion in time-share mode to digital data with a minimum 12-bit accuracy with respect to the applied analog input signals. The digitized data is supplied to an on-board processor 23 having Electrically Erasable Programmable Read-Only Memory (EEPROM) 24 with storage locations therein for storing the calibration data for the sensors, as later described herein. The processor 23 also includes a frequency compensation network 26 for further manipulating the sensor outputs, as described below. One suitable processor 23 is the DSP processor Model TMS 320C50 available from Texas Instruments, Inc. of Dallas, Tex.

The on-board processor 23 may be controlled to perform various calibration and operational routines via the conventional RS-232 controller port 25. The processor 23 may supply output data via a Digital-to-Analog (D/A) converter 27 for analog outputs per sensor in time-shared mode, or may provide output data per sensor as pulse-width modulated (PWM) output signal 29 in time-shared mode.

As illustrated in the flow chart of FIG. 3, data from all of the sensors 9-11, 13-15, and 17 (and 18 a-18 c, optionally) (FIG. 2) in one processing cycle are converted 31 in time-sequenced, shared mode by A/D converter 21 for storage in selected memory locations of the EEPROM 24. This digital data is converted 33 by the processor 23 to the sensed variables of accelerations and angular rates of the sensors within the assembly relative to the respective X, Y, and Z axes. This step is done using the calibration data stored in the EEPROM via application of the Sensor Compensation formulas, as set forth in Appendix A. Appendix A to Appendix G are provided below. A method of determining the proper calibration data (coefficients) in the Sensor Compensation formulas is described in detail below with reference to FIG. 6. An implementing program in ‘C’ or assembly language may be prepared in conventional manner to control a processor 23 that can execute solutions to the Sensor Compensation formulas at 100 H_(z) or faster rates. A DSP processor Model TMS320C206 available from Texas Instruments and operating on program code written in ‘C’ is suitable for the purpose. As stated above, optional magnetic sensors aligned with each of the X, Y, and Z axes may also be used to stabilize heading or yaw in addition to roll and pitch. The acceleration and rate sensors may then be calibrated 35 using calculations of the calibration coefficients, as detailed later herein. FIG. 6 below illustrates a method of performing the initial or “factory” calibration for the attitude measurement sensor in accordance with the present invention.

The angular rate signals are then integrated into a quaternion representation of attitude. The quaternion update formulas, and normalization of the quaternion, detailed in Appendix C, are further discussed below with reference to FIG. 7. The quaternion update 37 is the preferred method of attitude update because of the simplicity of the formulas and the small number (four) of variables that must be computed. Note that the integration is a function of not only the sensed angular rate but also the corrective angular rate as defined by ωcx, ωcy, ωcz. The generation of the corrective angular rate terms are described below in the text that follows. The incorporation of corrective angular rates prevents long term drift and instability that would be caused by the use of rate sensors alone. After the quaternion is computed, it is normalized to have a magnitude of one (1).

Once the quaternion has been updated to reflect the instantaneous orientation of the platform or object, the quaternion is converted 39 to a direction cosine matrix in preparation for computing the corrective rate signals ωcx, ωcy, ωcz. The formulas for the direction cosine matrix are set forth in Appendix D. A direction cosine matrix (like the quaternion) also completely characterizes the attitude orientation of a body. The direction cosine matrix, also referred to as a rotation matrix, is in fact a representation of the three rotations about the defined three axis (X, Y, and Z) needed to rotate a body from a level orientation (relative to gravity), to the final orientation desired. Hence the relationships in Appendix D describe how the elements of the quaternion, which also describes such orientation, can be converted to the nine terms needed to define the direction cosine matrix. The variables in Appendix D then include the definition of the direction cosine matrix itself in the form of a 3 by 3 matrix (nine terms) dc[3][3], and the conversion of the four quaternion elements a, b, c and d into the direction cosine matrix.

The direction cosine matrix is used to convert the acceleration vector of the platform or object into level frame readings that indicate 41 the true acceleration of the platform without tilt, as set forth in Appendix B. If, while the unit is sitting statically, there is a sensed level frame acceleration, one of two things has occurred. The solution for the attitude of the platform or object has drifted due to rate sensor drift, or the platform is moving linearly and accelerating in level frame coordinates.

The level frame accelerations are used to generate a corrective rate signal 43. There are several different methods of generating corrective rate signals, including Kalman or other conventional adaptive filtering, fixed gain scheduling, or non-linear gain scheduling. The Kalman filter/adaptive approach is optimal but involves extreme complexity (and leads to a relatively larger-sized and more expensive device). The proportional gain scheduling and non-linear gain (fixed-rate gain) scheduling are efficient and accurate enough for most scenarios, as detailed in Appendix E. For a setting of proportional gain, the corrective rate signals ωcx is obtained by multiplication of the level frame acceleration variable alev[2] (obtained during factory calibration) with the variable KG. The KG value can be considered a gain representing the magnitude of the correction, is user selectable and is described below. For a setting of non-linear, or fixed-rate gain, the corrective rate signal ωcx is obtained by multiplication of the factor (−1) with the variable UG for alev[2]>0.0. The UG value can be considered a gain representing the magnitude of the fixed-rate correction, is also user selectable and is described below. Additionally, FIG. 5A shows the plot of error correction for proportional gain schedule and FIG. 5B shows the plot of error correction for non-linear gain schedule.

As a further option, the gain amount for the correction factors may also be adjusted by the user of the system of the present invention. This option permits the user to modify the system output for various reasons such as factors in the environment of the system, noise limitations, stability criteria, and the like. An example for making gain correction user selectable is to allow for the possibility of providing useful data during a rapidly maneuvering mission. There is a tradeoff between how much error in the gyros the algorithm can overcome with a low gain correction, compared to the errors induced from having a high gain correction while experiencing large maneuvering accelerations. If the user has knowledge of the intensity of upcoming maneuvers or complete control of the flight profile, then an adapted gain correction scheme can be developed by minimizing the gain correction during the high acceleration portions, and increasing the gain correction when not accelerating.

As further shown in FIG. 3, a corrective rate for the Z (yaw) axis acceleration may be generated 45 based upon the measurements of the magnetic sensors 18 a-18 c, as shown in FIG. 2. Regarding gyroscopic errors attributable to heading or directional deviations, a GPS receiver can be used to measure heading of a platform that is moving and that supports the assembly of sensors 9-11, 13-15, and 17. Another way to measure heading is to use magnetic sensors to measure Earth's magnetic field in the same assembly of the rate sensors and accelerometers. The heading thus measured can optionally be used to stabilize the yaw axis from drift. This capability yields a directional gyro measurement without any additional cost. The formulas for stabilizing heading are detailed in Appendix F.

Although the attitude solution is computed and stored internally as a quaternion and direction cosines matrix, it is most conveniently transmitted in Euler Angle format which is chosen because of its small size (3 variables versus 4 for quaternion and 9 for direction cosines matrix) and because it is interpreted as a ‘real’ angle about an axis. The Euler Angles are extracted 47 from the direction cosines matrix, as detailed in Appendix G, and are supplied via the interface 25 to the RS 232 bus.

Thereafter, temperature corrections, and other corrections, can be digitally incorporated into the output data using correction values derived and stored in look-up tables in conventional manner. Specifically, for temperature calibration, the entire assembly may be operated at selected elevated temperatures to store acceleration and angular rate data at storage locations indexed by temperature values, and such data with associated corrections for temperature may thereafter be accessed from storage locations identified by the sensed operating temperature.

Similarly, look-up table corrections may also be prepared for operation in particular applications such as conventional camera stabilization platforms in which directional misalignments and non-linearities may be prepared in a look-up table indexed, for example, by angular orientations.

One-time factory calibration of the entire assembly of accelerometers and angular rate sensors and temperature sensor is typically required to correct for non-linearities of response, misalignments relative to the coordinate axes, and the like. Specifically, conventional accelerometers commonly produce an output linearly proportional to the input acceleration, with an offset value. Thus: Voltage out=Scale Factor*Acceleration+Offset  (Eq. 1)

For calibration, known accelerations are applied in axial alignment in order to compute the scale factor and the offset from the resulting output voltages. Gravity along the Z axis provides a convenient reference, but since minor variations occur in gravity, it is important to determine gravity at the site of the calibration, and this can be accomplished very precisely by referencing standard formulas and handbooks that contain the exact gravitational constant for every longitude and latitude on Earth. A level surface on X-Y plane provides a convenient reference of zero (0) acceleration, thereby allowing determination of the offset voltage (also known as “bias”).

Similarly, conventional angular rate sensors commonly produce an output voltage that is linearly proportional to the input angular rate, plus an offset. Thus: Voltage out=Scale Factor*Angular Rate+Offset  (Eq. 2)

To calibrate such angular rate sensor, the sensor offset may be measured as an output voltage while the sensor is not moving (neglecting Earth's rotation as not significantly affecting the offset results). However, measuring scale factor traditionally requires an elaborate rotational table to subject the assembly to fixed angular rate for producing a resultant output voltage. Alternatively, in accordance with the present invention, from Equation 2, above: V out−Offset=Scale Factor*Rate  (Eq. 3) ∫(V out−Offset)dt=Scale Factor*∫(Rate)dt  (Eq. 4) ∫(V out−Offset)dt=Scale Factor*Angle  (Eq. 5)

Equations 3 and 4 above describe algebraic and linear mathematical operations on Equation 2, namely the subtracting of both sides of Equation 2 by the offset, and then performing the integration operator on both sides of Equation 4. Equation 5 then defines the notion that the integral of the angular rate is in fact the angle. Since all variables of Equation 5 are determined except for scale factor, this parameter of a sensor can therefore be conveniently determined and used in the processing to solve for angular rate, given a sensor voltage, as detailed in Appendix A.

Regarding accelerometer alignment errors, these errors represent cross coupling between the axes of sensitivity attributable to misalignment of an accelerometer with the associated coordinate axis of responsiveness. Of course, if each accelerometer can be precisely aligned with its associated coordinate axis, then misalignment error is eliminated. However, machining tolerances and fabrication anomalies contribute to unpredictable misalignment errors, and accordingly, cross axis calibration following assembly is employed to improve accuracy of acceleration responses. Specifically, the assembly of sensors is placed on each of its three axes and an output is recorded. The value of the output is subtracted from the true input acceleration which will be zero on two axes and 1G on the axis exposed to gravitational field. The resulting data is organized into a matrix of 9 elements. This matrix is inverted in conventional manner and the result is a compensation matrix which converts measurements that have cross-axis sensitivities to true accelerations.

FIG. 6 illustrates a method of obtaining and setting the correction factors described above. The procedure for obtaining the correction factors will hereafter be referred to as “the calibration procedure.” The calibration procedure is designed to adaptively estimate the correction factors for the six sensors in question. Optional magnetometer calibration is generated by taking measurements in a Helmhotz Coil. Calibrating a complicated six-axis system is a difficult prospect when considering the amount of errors that are inherently part of the measurement technology employed by the accelerometers and gyros. The difficulty lies in the fact that to estimate the error factors in any calibration technique requires understanding the underlying properties of each error to generate data that reflects the error specifically, and seldom are the errors uncoupled enough to isolate each separate error source with much confidence.

The procedure developed provides a technique which estimates all the error parameters at once from a single set of data, and generates the proper compensation for each error source. The technique employs an adaptive filtering scheme, a Kalman Filter, which processes a set of accelerometer and gyro readings from a predefined set of maneuvers. In essence, the calibration involves obtaining data from the sensors as the system 100 is placed on a leveled table 105, rotated about each axis and laid down on each face of the cube enclosing the system 100, and then processing the data with the Kalman Filter software which generates the compensation tables. As a final step the calibration compensation parameters are loaded into the EEPROM 24, from which the DSP 23 of FIG. 2 is able to obtain the parameters to apply the compensation to the raw accelerometer and gyro measurements to achieve calibrated data. The Kalman filter is a tried and true method of using a computer processor to estimate a set of parameters from a set of measurement data. The measurement data can be a direct measurement of the parameter, also known as a state, or a measurement of a signal that in some way has a mathematical relationship to the state the filter is trying to estimate. Such filter structure is made up of two separate components including a state model and a measurement model. The state model is a detailed mathematical representation of the states, which is used to simulate their behavior and obtain a prediction of what values the states will have at some time in the future. The measurement model derives a correction to the predicted state based on the measurement data, and it is this corrected prediction of the state that is referred to as the final state estimate. In the calibration procedure Kalman Filter, the states that are estimated are the sensor correction factors or calibration parameters. A complex mathematical model of the behavior of the parameters and their interdependence makes up the state model. It uses the accelerometer and gyro data from the maneuvers to help in the prediction of the behavior of the parameters. The filter then infers from the maneuvers themselves information that it uses as a measurement of the parameters. For instance, the filter can determine when it has arrived at a stationary point in a maneuver, and therefore assumes that accelerometers should measure zero with one axis along the gravity axis, and that the gyros should also measure zero. This information is processed by the measurement model, which deems any gyro data or gravity axis offset at this point as a measurement of the parameters, and forms a correction for the predicted parameters from the state model. A list of the parameters currently estimated by the filter is represented in the Table 1 below. Each parameter is weighted for its impact on the overall performance of the filter. The marks shown below depict those parameters deemed important for the represented sensor.

TABLE 1 Gyros or Rate Sensors Accelerometers Bias X X Scale Factor X X Squared Non-Linearity X Misalignment X X

A Kalman filter algorithm for navigating the DMU in a local level frame during calibration is described above. More specifically, the compensation parameters can be determined using a calibration procedure designed to adaptively estimate the calibration parameters. Calibrating a complicated sensor like the DMU is a difficult prospect when considering the errors that are inherently part of the measurement technology employed by the accelerometers and rate sensors. Traditional methods of calibration involve generating enough data from rate and vibration tables and then using curve-fitting techniques to determine the correct compensation. The difficulty lies in the fact that to estimate the error factors in any calibration technique requires understanding the underlying properties of each error to generate data that reflects the error specifically, and seldom are the errors uncoupled enough to isolate each separate error source with much confidence.

Thus, utilizing an adaptive calibration technique based on a Kalman filter involves generating data from the DMU as it is placed on a leveled table, rotated about each axis and laid down on each face of the cube-shaped DMU package 100, as illustrated in FIG. 6, and then processing the data with the Kalman filter software to generate the compensation tables. As a final step the calibration compensation parameters are coded into the DMU's onboard processor and memory for application as compensation to the raw accelerometer and rate sensor measurements to achieve calibrated data.

In the Kalman filter that is applied during calibration, the states that are estimated are the calibration parameters and the reference measurements are the accelerometer and rate sensor data from the maneuvers and from known static positions of the packaged DMU 100 on the leveled table 105. The filter then infers from the maneuvers the information that it uses as a measurement of the parameters. For instance, the filter can determine when it has arrived at a stationary point in a maneuver, and therefore assumes that accelerometers should measure zero, except for the measure of 1 along the gravity axis, and that the rate sensors should also measure zero. This information is processed by the measurement model, which regards any variations from these conditions in the rate sensor data or gravity axis at this point as a measurement of the offset or bias parameters, and forms a correction for the predicted parameters from the state model. A list of the parameters estimated by the filter is represented in Table 1, above. Each parameter may be weighted for its impact on the overall performance of the filter. The marks shown in Table 1 depict those parameters deemed important for the represented sensor.

FIG. 7 illustrates a method of updating and normalizing a quaternion that is obtained from the sensor outputs. Appendix C defines the update and normalization procedures for the quaternions. The update portion is in fact a propagation of the quaternion vector as it propagates in time. In order to characterize how the quaternion changes in time, an equation is created which explicitly defines the time dependency of the quaternion (or its derivative), and this equation is referred to as a differential equation. The propagation is then obtained by calculating the solution to the differential equation. In order to solve the differential equation we need to integrate 150 the equation which then removes the time dependence of the derivative of the quaternion, and allows us to obtain the value of the quaternion at any time. In order to maintain complete stability of the calculation, one of the properties of the quaternion that must be maintained is that the magnitude (the square root of the sum of the squares) of the quaternion vector must always equal one (1). This is achieved by normalizing 37 the quaternions. The variables in Appendix C describe both the updating and normalization process. The quaternion is represented by a, b, c and d, and the angular rate vector (calibrated gyro measurements) is represented by ωc[3]. The four temporary terms a4, b4, c4 and d4 represent the derivative of the quaternion, and the four equations for these terms represent the differential equation for the quaternion vector. Notice the dependence of the derivative (time rate of change) of the quaternion on the angular rate terms which really represent the rate of change of the rotation about each axis X, Y, and Z. Also notice that the corrective angular rates ωcx, ωcy and ωcz are also present in the differential equation. This is in effect how the angular rate terms obtained from the gyros are corrected. The update quaternion section and the four equations using the quaternion terms define the integration of the differential equation process. The time dependency on the derivative of the quaternion is solved for, and therefore the quaternion vector itself is calculated. The final section then normalizes the calculated quaternion thereby assuring that the magnitude of the quaternion will always be one (1).

Reference is now made to FIGS. 4A and 4B in order to discuss a further compensation process that may be provided by the system in accordance with the present invention. The bandwidth of conventional sensors is commonly too narrow (e.g. about 10 Hertz) for many applications requiring quick stabilization to produce accurate output data rapidly. In such applications, a frequency-compensating network 26, as shown in FIG. 4A in either digital or analog form, may be introduced into the circuit to operate on sensor output signals, and may include a differentiator 40 and summing junction 42 followed by a low pass filter 44. Specifically, the angular rate signal, c, is applied to differentiator 40 and to summing network 42 which is also connected to receive the output of the differentiator 40. A low-pass filter 44 having a bandwidth to about 100 Hertz receives the combined angular rate signal, ω, and the differentiated angular rate signal at the output of summing network 42 to provide the compensated angular rate signal, ωc, having higher frequency components and wider bandwidth, as shown in FIG. 4 b, than the initial angular rate signal.

Thus, the frequency compensation stage performs frequency compensation to the gyros and accelerometers which can provide enhanced dynamic response of, reduce the noise in, and reduce the sensitivity to vibration of the quaternion update. In other words, performing frequency compensation is performed to the gyro sensor data which expand the operational bandwidth of the gyros to provide updates to the quaternion under dynamic conditions which the gyro sensor alone would not be able to track, or which compress (filter) the gyro and accelerometer bandwidth to reduce noise and to reduce vibration sensitivity in the quaternion calculation.

As a further option, the user may turn off the low-pass filter 44 so that the above filter compensation technique is not performed.

Referring now to the block schematic diagram of FIG. 8, an additional slave co-processor 51 is included in the system to perform the Kalman filtering computation. As in the embodiment previously described with reference to FIG. 2, data acquisition components include three-axes gyros 53 and three-axes accelerometers 55, and optionally magnetic or compass or other heading references (not shown), together with temperature monitor 57 and an A/D converter 59 under control of the main or master processor 61 that includes non-volatile memory for storing calibration error correction data for the data acquisition components, all in a manner as previously described herein. The main processor 61 performs the attitude computation, as previously described herein, and also performs system control monitoring. The computed data or raw sensor data in digital form may be accessed through a serial communication bus (e.g., RS232) 53, as previously described herein, or may be accessed in analog form with error compensation included via a D/A converter 65 in the analog output channel 67.

In order to run the Kalman filter efficiently, a second or slave co-processor 69 is closely coupled to the main processor 61 and is used to optimally implement the necessary algorithms, as described in the enhanced implementation data herein. As illustrated in FIG. 9, and as previously described herein, data in the process flows from sensor array through a compensation stage, and then an attitude computation stage.

At each point in the process, the sensor outputs are processed to produce optimum performance depending upon the application and temperature and other environmental conditions. The optimizing parameters are determined during manufacturing and calibration and are permanently stored in an EEPROM, as previously described herein.

In accordance with this embodiment of the present invention, the attitude determination algorithm is divided into two separate entities. Information about angular rate as measured by rate sensors is integrated in time in an attitude processor routine. If the initial attitude of the vehicle was known exactly and if the rate sensors provided perfect readings then the attitude processing would suffice. However, the initial attitude is seldom known, and rate sensors typically provide corrupted data due to bias drift and turn-on instability. Without an adaptive filter structure such as a Kalman filter and separate independent measurements, the computed navigation results would diverge off the true trajectory. The Kalman filter attitude-correction routine therefore provides an on-the-fly calibration by providing corrective signals (referred to as correction quaternion terms) to the computed attitude processor quaternion and a characterization of the rate sensor bias state, with the accelerometers providing an attitude reference from gravity.

Referring now to FIG. 10, the reference plane described above with respect to FIG. 1 may be considered as a coordinate frame for the attitude measurement. The body axis of a vehicle such as an aircraft is defined as the coordinate frame with positive x through the vehicle nose, positive y through the right wing, and positive z down to complete the right-handed orientation of three axes. Its origin is nominally located at the vehicle center of gravity (CG). In FIG. 10, the body frame of the vehicle is shown relative to the tangent frame or local level horizontal frame. In this construct, the body axis 71 is chosen to point toward north along its x-axis when there is no yaw angle. Therefore when the vehicle attitude is zero, or that the Euler angles of roll, pitch, and yaw are zero, the transformation from body frame to tangent frame is simply:

${{CB}\; 2\; T} = \begin{bmatrix} 1 & 0 & 0 \\ 0 & 1 & 0 \\ 0 & 0 & 1 \end{bmatrix}$

Here the matrix represents the “cosine rotation matrix which converts from body (2) to tangent frame”. The term tangent frame can be used interchangeably, with the term level frame as used in the previous description. This serves as the starting point for further rotation of the body in the tangent frame due to changes in vehicle attitude. Several angles defined in the FIG. 10 are of importance for the vehicle. The centerline of the vehicle 73 is shown displaced from the vehicle's velocity vector 75 in the tangent frame. The angles which the velocity vector 75 makes with respect to the vehicle centerline 73, are the typical aerodynamic control angles, including angle of attack: α, and angle of sideslip β. The angles that the velocity vector makes with respect to the tangential plane are the typical air velocity angles including flight path angle λ and heading angle γ. The Euler body angles, which the centerline of the vehicle body 73 makes with respect to the tangential frame are the pitch θ and yaw ψ angles. The vehicle body roll angle φ is rotated along its centerline. The Euler angles describe the vehicle attitude and form a 3-2-1 rotation of the body in the tangent frame. In explicit terms the rotation matrix is:

$\begin{matrix} \begin{matrix} {{{CB}\; 2T} = {{{\begin{bmatrix} 1 & 0 & 0 \\ 0 & 1 & 0 \\ 0 & 0 & 1 \end{bmatrix}\begin{bmatrix} {c\;\psi} & {{- s}\;\psi} & 0 \\ {{s\;\psi}\;} & {c\;\psi} & 0 \\ 0 & 0 & 1 \end{bmatrix}}\begin{bmatrix} {c\;\theta} & 0 & {s\;\theta} \\ 0 & 1 & 0 \\ {{- s}\;\theta} & 0 & {c\;\theta} \end{bmatrix}}\begin{bmatrix} 1 & 0 & 0 \\ 0 & {c\;\phi} & {{- s}\;\phi} \\ 0 & {s\;\phi} & {c\;\phi} \end{bmatrix}}} \\ {{{CB}\; 2T} = \begin{bmatrix} {c\;\psi\; c\;\theta} & {{{- s}\;\psi\; c\;\phi} + {c\;\psi\; s\;\theta\; s\;\phi}} & {{s\;\psi\; s\;\theta} + {c\;\psi\; s\;\theta\; c\;\phi}} \\ {s\;\psi\; c\;\theta} & {{c\;\psi\; c\;\phi} + {s\;\psi\; s\;\theta\; s\;\phi}} & {{c\;\psi\; s\;\phi} + {s\;\psi\; s\;\theta\; c\;\phi}} \\ {{- s}\;\theta} & {c\;{\theta s\phi}} & {c\;\theta\; c\;\phi} \end{bmatrix}} \end{matrix} & \left( {{Eq}.\mspace{14mu} 7} \right) \end{matrix}$

-   -   where c is abbreviation for cosine; and         -   s is abbreviation for sine.

From this rotation matrix which will transform a vector from the body frame into the tangent frame, the attitude Euler angles can be derived as follows:

$\begin{matrix} \begin{matrix} {\phi_{({roll})} = {a\;{\tan\left( \frac{{CB}\; 2{T\left( {3,2} \right)}}{{CB}\; 2{T\left( {3,3} \right)}} \right)}}} \\ {\theta_{({pitch})} = {{- a}\;{\sin\left( {{CB}\; 2{T\left( {3,1} \right)}} \right)}}} \\ {\psi_{({yaw})} = {a\;{{\tan\left( \frac{{CB}\; 2{T\left( {2,1} \right)}}{{CB}\; 2{T\left( {1,1} \right)}} \right)}.}}} \end{matrix} & \left( {{Eq}.\mspace{14mu} 8} \right) \end{matrix}$

As previously described herein the attitude estimation algorithm processed provides stable Euler roll, pitch angles. These angles are determined by integrating the rate signals into a quaternion representation of attitude (or the CB2T matrix). The quaternion formulation for the transformation is repeated below. Following Euler's theorem, the quaternion is a representation of a rotation about an axis of rotation (e₁, e₂, and e₃) by an angle φ. The components of the quaternion are:

$\begin{matrix} \begin{matrix} {\overset{\_}{q} = {\begin{bmatrix} q_{1} \\ q_{2} \\ q_{3} \end{bmatrix} = \begin{bmatrix} {{\sin\left( \frac{\varphi}{2} \right)}{\mathbb{e}}_{1}} \\ {{\sin\left( \frac{\varphi}{2} \right)}{\mathbb{e}}_{2}} \\ {{\sin\left( \frac{\varphi}{2} \right)}{\mathbb{e}}_{3}} \end{bmatrix}}} \\ {q = \begin{bmatrix} q_{0} \\ \overset{\_}{q} \end{bmatrix}} \\ {q_{0} = {\sqrt{1 - {{\overset{\_}{q}}^{T\;}\overset{\_}{q}}} = {\cos\left( \frac{\varphi}{2} \right)}}} \end{matrix} & \left( {{Eq}.\mspace{14mu} 9} \right) \end{matrix}$

The quaternion vector component representing the axis of rotation is q, and the quaternion scalar component q₁ represents the angle of rotation. The cosine rotation matrix is directly defined by the quaternion as:

$\begin{matrix} {{{CB}\; 2\; T} = \begin{bmatrix} {q_{0}^{2} + q_{1}^{2} - q_{2}^{2} - q_{3}^{2}} & {2\left( {{q_{1}q_{2}} - {q_{0}q_{3}}} \right)} & {2\left( {{q_{1}q_{3}} + {q_{0}q_{2}}} \right)} \\ {2\left( {{q_{1}q_{2}} + {q_{0}q_{3}}} \right)} & {q_{0}^{2} - q_{1}^{2} + q_{2}^{2} - q_{3}^{2}} & {2\left( {{q_{2}q_{3}} - {q_{0}q_{1}}} \right)} \\ {2\left( {{q_{1}q_{3}} - {q_{0}q_{2}}} \right)} & {2\left( {{q_{2}q_{3}} + {q_{0}q_{1}}} \right)} & {q_{0}^{2} - q_{1}^{2} - q_{2}^{2} + q_{3}^{2}} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 10} \right) \end{matrix}$

In this way, the quaternion that makes the transformation is:

$\begin{matrix} {{{QB}\; 2T} = \begin{bmatrix} q_{0} \\ q_{1} \\ q_{2} \\ q_{3} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 11} \right) \end{matrix}$

Finally the body attitude is calculated from the QB2T quaternion (body to tangent) by employing the derivative of the quaternion formulation described below:

$\begin{matrix} {\lambda = {\left\lbrack {{QB}\; 2T} \right\rbrack = \left\lbrack {\frac{1}{2}*\Omega_{{Bodyrate}\;}*{QB}\; 2T} \right\rbrack}} & \left( {{Eq}.\mspace{14mu} 12} \right) \end{matrix}$

The quaternion equation contains a matrix representation Q of the angular rate of change of the coordinate frame in question. The matrix is made up of the angular rates about each coordinate axis:

$\begin{matrix} {{\Omega = \begin{bmatrix} 0 & {- \omega_{x}} & {- \omega_{y}} & {- \omega_{z}} \\ \omega_{x} & 0 & \omega_{z} & {- \omega_{y}} \\ \omega_{y} & {- \omega_{z}} & 0 & \omega_{x} \\ \omega_{z} & \omega_{y} & {- \omega_{x}} & 0 \end{bmatrix}}{\overset{\_}{\varpi} = {\begin{bmatrix} \omega_{x} \\ \omega_{y} \\ \omega_{z} \end{bmatrix}\begin{matrix} {{Angular}\mspace{14mu}{rate}\mspace{14mu}{about}\mspace{14mu}{the}\mspace{14mu} X\text{-}{axis}} \\ {{Angular}\mspace{14mu}{rate}\mspace{14mu}{about}\mspace{14mu}{the}\mspace{14mu} Y\text{-}{axis}} \\ {{Angular}\mspace{14mu}{rate}\mspace{14mu}{about}\mspace{14mu}{the}\mspace{14mu} Z\text{-}{axis}} \end{matrix}}}} & \left( {{Eq}.\mspace{14mu} 13} \right) \end{matrix}$

The solid-state gyros sense the body angular rates and the differential equation above is integrated to obtain the propagated quaternion QB2T. The relationships described above then provide the cosine rotation matrix from the quaternion and finally the attitude angles of roll, pitch and yaw from the cosine rotation matrix.

As previously described herein, a Kalman filter uses acceleration information, in particular the level (or tangent) frame acceleration information, to generate a corrective rate signal, thereby removing drift and improving accuracy of the attitude measurement. In another embodiment of the present invention, the attitude correction by the Kalman filtering achieves improved performance due to its ability to estimate the attitude errors and rate sensor bias (offset) states. In this embodiment, an absolute attitude error estimate is provided to the trajectory to correct any errors due to physical noise disturbances and rate sensor errors, as well as a characterization and “tracking” of the rate sensor biases which in effect provide an online rate sensor calibration. The filter model in this embodiment is an extended Kalman filter formulation made up of a linearized attitude error and rate sensor bias state model, and a nonlinear attitude quaternion error measurement model. The state model predicts where the attitude errors and rate sensor bias states will propagate based on input data from the rate sensors, and the measurement model corrects this prediction with the real world attitude error measurements obtained from the accelerometer gravity reference (also referred to as level frame acceleration), and from the leveled magnetometer heading reference. This balance of state modeling with real world parameters gives the Kalman filter the adaptive intelligence to assign appropriate confidence levels on its two components.

In this embodiment, the Kalman filter is designed to correct the trajectory calculated by the attitude processor 61 and its state space is confined to estimating errors or perturbations in that attitude trajectory due to corrupt sensors. This is referred to as generating a trajectory perturbation state vector which includes attitude perturbations and sensor characterization that model the absolute error sources in the sensors, composed mainly of the rate sensor biases, or offsets.

The attitude perturbation is defined to be the error in the attitude processor knowledge of the body attitude with respect to the tangent frame. The filter state elements and their sizes are defined as follows:

$\begin{matrix} {{\delta\;{\hat{x}}_{est}} = {\begin{bmatrix} {\delta\;\overset{\_}{q}} \\ {\delta\; g_{b}} \end{bmatrix}\begin{matrix} \,_{3 \times 1} \\ \;_{3 \times 1} \end{matrix}}} & \left( {{Eq}.\mspace{14mu} 14} \right) \end{matrix}$

There are three rate sensor bias estimates δg_(b) for the rate sensors on each axis in the vehicle body frame. The attitude perturbation is modeled as a quaternion and is similar to Eq. 9. It defines the perturbation in vehicle attitude and is used to update the body-to-tangent frame cosine rotation matrix CB2T, thus providing a means to correct or “rotate” the current body frame to the latest estimate for the body frame.

$\begin{matrix} {{\delta\;\overset{\_}{q}} = {{\begin{bmatrix} {\delta\; q_{1}} \\ {\delta\; q_{2}} \\ {\delta\; q_{3}} \end{bmatrix}\mspace{31mu}\delta\; q} = {{\begin{bmatrix} {\delta\; q_{0}} \\ {\delta\; q_{1}} \\ {\delta\; q_{2}} \\ {\delta\; q_{3}} \end{bmatrix}\mspace{31mu}\delta\; q_{0}} = \sqrt{1 - {\delta\;{\overset{\_}{q}}^{T}\delta\;\overset{\_}{q}}}}}} & \left( {{Eq}.\mspace{14mu} 15} \right) \end{matrix}$

In presenting the state transition matrix below, the matrix cross product formulation is employed throughout. The definition of the notation is as follows:

$\begin{matrix} {{\overset{\_}{u} \times \overset{\_}{v}} = {{\left\lbrack {\overset{\_}{u} \times} \right\rbrack\overset{\_}{v}} = {\begin{bmatrix} 0 & {- u_{z}} & u_{y} \\ u_{z} & 0 & {- u_{x}} \\ {- u_{y}} & u_{x} & 0 \end{bmatrix}\begin{bmatrix} v_{x} \\ v_{y} \\ v_{z} \end{bmatrix}}}} & \left( {{Eq}.\mspace{14mu} 16} \right) \end{matrix}$

The attitude perturbation model contains most of the dynamical information, and therefore the attitude error reference which is obtained from the accelerometers and which provides a clear measure of the vehicle attitude in the tangent frame is significant. The rate sensor signals are used directly in the state transition matrix making it a time-varying process, as well as making it sensitive to the quality of the sensor signals. Very noisy rate sensor measurements should be pre-filtered, as previously discussed herein, before introducing them into the system, especially if that noise is electronic or high-frequency vibration disturbances above the bandwidth of the vehicle performance. The matrix is presented in the relationship below:

$\begin{matrix} {{{\delta\;{\overset{.}{\hat{x}}}_{est}} = {{A_{state}\delta\; x_{est}} + Q}}{{\delta\;{\overset{.}{\hat{x}}}_{est}} = {\begin{bmatrix} {\delta\;\overset{.}{\overset{\_}{q}}} \\ {\delta\;{\overset{.}{g}}_{b}} \end{bmatrix} = {{\begin{bmatrix} A_{qq} & A_{qe} \\ 0_{3 \times 3} & 0_{3 \times 3} \end{bmatrix}\begin{bmatrix} {\delta\;\overset{\_}{q}} \\ {\delta\; g_{b}} \end{bmatrix}} + \begin{bmatrix} \omega_{\overset{\_}{q}} \\ \omega_{g_{b}} \end{bmatrix}}}}} & \left( {{Eq}.\mspace{14mu} 17} \right) \end{matrix}$

From the perturbation state dynamics defined above, certain clear relationships are formed. The attitude perturbation δ q dynamics are affected by errors due to coupled sensors in the rate sensor, with absolute errors in attitude that explain its dependency on the rate sensor measurements as well as the rate sensor bias terms. Each term is defined below: A _(qq)=Gyro_(Body) *δ q ^(T)*Gyro_(Body)−[(Gyro_(Body)+0.5*(2*δ q ×Gyro_(Body) +* g _(b)))×]A _(qe)=0.5*I ₃ −[δ q×]  (Eq. 18)

Using a quaternion formulation for attitude perturbations provides the advantage of using the higher order terms of the quaternion, and improved dynamic behavior of the quaternion. Perturbations in Euler angles, and its dynamic propagation is a very simple first order approximation that breaks down if the attitude errors grow large. The state process noise terms ω defined in the state dynamic equations (Eq. 17) are modeled as white noise for all the states. The noise covariance matrix for the state transition noise terms is labeled Q and is defined as a diagonal 6×6 matrix with values initially chosen to achieve the desired filter performance from flight trajectory simulation.

In order to improve the attitude error estimation portion of the Kalman filter, an adaptive component was added to the state model noise covariance which allowed the filter to respond very quickly to situations in which the reference information is probably corrupted. Two dynamic conditions cause the accelerometer reference of gravity to be corrupted, including:

1. Dynamic acceleration changes due to change-in-velocity maneuvers; and

2. Coordinated Turn Maneuvers (or turns generating significant centripetal acceleration).

In the first condition, the accelerometers measure the true body acceleration due to a change-in-velocity, which will corrupt its measurement of gravity and can lead to a larger than true attitude reference. In the second condition, the accelerometers measure the combined (null) effect of gravity and centripetal acceleration, which leads to a smaller than true attitude reference. The goal then is to determine when these situations arise and to provide the proper adaptive change to the state model noise covariance. The two components that make up this model are a dynamic maneuver determination test, and a coordinated turn determination test, as illustrated in the flow charts of FIGS. 11 and 12. The dynamic maneuver determination test is based upon the acceleration data obtained from the accelerometers. As defined in the flow diagram of FIG. 11, the three vector accelerations 81 are converted into a lateral/longitudinal magnitude of acceleration term 83 which excludes the Z-acceleration component. This magnitude signal is then passed through a high-pass filter 85 to remove any bias in the signal. The resultant signal provides a measure of the amount of “maneuvering” acceleration sensed by the accelerometers in the X-Y plane. This is the plane of reference used to obtain the attitude with respect to gravity information used by the Kalman filter. The signal is then checked against a threshold value 87 and, if in excess of the threshold value 89, the algorithm assumes that the vehicle is maneuvering and will no longer accept the attitude computation as correct with respect to gravity reference.

The coordinated turn maneuvers test is based solely on the yaw gyro signal 91 which is first passed through low-pass filter 93, as shown in FIG. 12, to remove typical yaw turn perturbations due to small flight or body corrections. The signal is then checked against a threshold 95 and, if in excess of the threshold 97, the algorithm assumes the vehicle is in a coordinated turn 99 or other turn maneuver that generates significant centripetal force. The algorithm accordingly lowers the state model noise covariance, which effectively lowers the gain and response of the Kalman filter. With the Kalman filter in a low-gain mode, attitude error build-up during a turn is kept to a minimum by maintaining those gyro bias estimates that were produced prior to the turn maneuver, and lowering the weighting on the accelerometer attitude reference which would otherwise attempt to force the attitude indication toward level.

The measurement model for the filter contains components that are nonlinear in nature. The attitude reference error measurements are direct measurements of the Euler angle errors, and are therefore a nonlinear combination of the quaternion perturbation states. They are obtained by rotating the body measured accelerometer signals into the tangent or level frame, and then calculating the attitude reference error by observing any residual non-level acceleration terms in the tangent and assigning the attitude error measurements based on the magnitude of the residual terms.

The heading reference error is obtained by calculating the heading direction as measured from the leveled magnetometers, and comparing this heading to the current calculated yaw angle obtained from the attitude trajectory that is determined from the integrated quaternion. The heading error measurement then is based on the magnitude of the residual angle error difference between the magnetometer heading and the calculated yaw. The following relationship describes the Kalman filter measurement model:

The reference residuals comprise the body accelerometer and

$\begin{matrix} {y_{meas} = {\begin{bmatrix} {\delta\;{roll}_{ref}} \\ {\delta\;{pitch}_{ref}} \\ {\delta\;{yaw}_{ref}} \end{bmatrix} - {\quad{\begin{bmatrix} {\delta\;{roll}_{est}} \\ {\delta\;{pitch}_{est}} \\ {\delta\;{yaw}_{est}} \end{bmatrix} = {{\begin{bmatrix} {ACCY}_{{TAN}\mspace{11mu}{residual}} \\ {ACCX}_{{TAN}\mspace{11mu}{residual}} \\ {Heading}_{residual} \end{bmatrix} - {\begin{bmatrix} {f_{1}\left( {\delta\; q} \right)} \\ {f_{2}\left( {\delta\; q} \right)} \\ {f_{3}\left( {\delta\; q} \right)} \end{bmatrix}\mspace{79mu} y_{meas}}} = {{{C_{meas}*\delta\; x_{est}} + {R_{meas}\mspace{20mu} y_{meas}}} = {{C_{meas}*\begin{bmatrix} {\delta\;\overset{\_}{q}} \\ g_{b} \end{bmatrix}} + \begin{bmatrix} G_{\delta\;\overset{\_}{q}} \\ G_{g_{b}} \end{bmatrix}}}}}}}} & \left( {{Eq}.\mspace{14mu} 19} \right) \end{matrix}$ magnetometer data and are obtained from the following relationship:

$\begin{matrix} {\mspace{79mu}{{{ACC}_{TAN} = {{{CB}\; 2T*{{ACC}_{BODY}\begin{bmatrix} {ACCX}_{{TAN}\mspace{11mu}{residual}} \\ {ACCY}_{{TAN}\mspace{11mu}{residual}} \\ {Heading}_{residual} \end{bmatrix}}} = \begin{bmatrix} {{{sign}\left( {ACC}_{{TAN}\; X} \right)}*\theta_{({ADAPT})}} \\ {{- {{sign}\left( {ACC}_{{TAN}\; Y} \right)}}*\phi_{({ADAPT})}} \\ {{{sign}\left( {Heading}_{ERR} \right)}*\psi_{({ADAPT})}} \end{bmatrix}}}\mspace{79mu}{{Heading}_{ERR} = {\psi_{({yaw})} - {Heading}_{Mag}}}\mspace{20mu}{{Heading}_{Mag} = {{a\;\tan\; 2{\left( {{MAGY}_{TAN},{MAGX}_{TAN}} \right)\begin{bmatrix} {MAGX}_{TAN} \\ {MAGY}_{TAN} \end{bmatrix}}} = {\quad\begin{bmatrix} {{{\cos(\theta)}*{MAG}_{X}} + {{\sin(\theta)}*{\sin(\phi)}*{MAG}_{Y}} + {{\cos(\phi)}*{MAG}_{Z}}} \\ {{{\sin(\phi)}*{MAG}_{Z}} - {{\cos(\phi)}*{MAG}_{Y}}} \end{bmatrix}}}}}} & \left( {{Eq}.\mspace{14mu} 20} \right) \end{matrix}$

The angle perturbation estimate functions represent the attitude error that the Kalman filter has estimated up to that point, and are obtained from the following relationship:

$\begin{matrix} {{{\tan\; 1} = {2.0*\left( {{\delta\; q_{2}*\delta\; q_{3}} + {\delta\; q_{1}*\delta\; q_{0}}} \right)}}{{\tan\; 2} = {1.0 - {2.0*\left( {{\delta\; q_{2}*\delta\; q_{2}} + {\delta\; q_{1}*\delta\; q_{1}}} \right)}}}{{\tan\; 3} = {2.0*\left( {{\delta\; q_{1}*\delta\; q_{2}} + {\delta\; q_{3}*\delta\; q_{0}}} \right)}}{{\tan\; 4} = {{1.0 - {2.0*{\left( {{\delta\; q_{2}*\delta\; q_{2}} + {\delta\; q_{3}*\delta\; q_{3}}} \right)\begin{bmatrix} {f_{1}\left( {\delta\; q} \right)} \\ {f_{2}\left( {\delta\; q} \right)} \\ {f_{3}\left( {\delta\; q} \right)} \end{bmatrix}}}} = \begin{bmatrix} {a\;\tan\; 2\left( {{\tan\; 1},{\tan\; 2}} \right)} \\ {a\;{\sin\left( {2.0*\left( {{\delta\; q_{0}*\delta\; q_{2}} - {\delta\; q_{1}*\delta\; q_{3}}} \right)} \right)}} \\ {a\;\tan\; 2\left( {{\tan\; 3},{\tan\; 4}} \right)} \end{bmatrix}}}} & \left( {{Eq}.\mspace{14mu} 21} \right) \end{matrix}$

The measurement matrix C_(meas) in Eq. 19 is calculated as:

$\begin{matrix} {C_{meas} = \begin{bmatrix} {{2*\delta\; q_{0}} - \frac{2*\delta\; q_{1}^{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{3}} - \frac{2*\delta\; q_{1}*\delta\; q_{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{2}} - \frac{2*\delta\; q_{1}*\delta\; q_{3}}{\delta\; q_{0}}} & 0_{1 \times 3} \\ {{{- 2}*\delta\; q_{3}} - \frac{2*\delta\; q_{1}*\delta\; q_{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{0}} - \frac{2*\delta\; q_{2}^{2}}{\delta\; q_{0}}} & {{{- 2}*\delta\; q_{1}} - \frac{2*\delta\; q_{2}*\delta\; q_{3}}{\delta\; q_{0}}} & 0_{1 \times 3} \\ {{{- 2}*\delta\; q_{3}} - \frac{2*\delta\; q_{2}*\delta\; q_{4}}{\delta\; q_{1}}} & {{{- 2}*\delta\; q_{2}} - \frac{2*\delta\; q_{3}*\delta\; q_{4}}{\delta\; q_{1}}} & {{{- 2}*\delta\; q_{1}} - \frac{2*\delta\; q_{4}*\delta\; q_{4}}{\delta\; q_{1}}} & 0_{1 \times 3} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 22} \right) \end{matrix}$ and is the linearized matrix representation that essentially transforms the Kalman filter estimated quaternion perturbation into the Kalman filter measurement attitude reference error.

Measurement noise covariances are defined from the performance of the accelerometers and magnetometers and are contained in R_(meas) in Eq. 19.

A conventional Kalman filter is employed and its function and typical nomenclature for coefficients, and the like, are described below. The filter state and transition matrix is first discretized, and then the discrete time Kalman filter is employed. Since the measurements come in at varying sample rate, a varying-rate filter configuration is employed.

During an update, the full Kalman filter is calculated which includes the prediction and correction steps. The equations follow: A _(k)=(I+Δt*A _(state)) δ x _(pred) =A _(k) *δ{circumflex over (x)} _(est) H=A _(k) *P _(est) *A _(k) ^(T) +Q _(k) K=H*C _(meas) ^(T)*(C _(meas) *H*C _(meas) ^(T) +R _(meas))⁻¹. P _(est)=(I−K*C _(meas))*H υ=(y _(meas) −C _(meas) *δ x _(pred)) δ{circumflex over (x)} _(est) =δ{circumflex over (x)} _(pred) +K*υ  (Eq. 23)

The measurement matrix C_(meas) is defined above in Eq. 22, and the state transition matrix A_(state) is defined in Eqs. 17 and 18, and the measurement noise covariance R_(meas) is defined above in Eq. 19. The measurement vector y_(meas) is defined from the attitude reference error calculation described in the measurement model discussion above and is represented in Eq. 19. The state process noise covariance Qk is a discretized form of the continuous state process noise covariance Q to account for the varying filter sample rate. Each element of the Kalman filter equations of Eq. 23 have been defined previously, and the interim terms such as H, and K and P_(est) are conventional in classic Kalman filter terminology.

In an alternative embodiment, an external velocity or airspeed reference may be used to aid in the determination of attitude. In order to improve roll, pitch, and heading performance during certain maneuvers, an external velocity aiding reference is incorporated into the attitude prediction algorithm. In situations where long sustained accelerations arise from the dynamics (as is possible in the distinct class of high performance aircraft), the algorithm may not be responsive enough, nor designed to handle long continuous changes in velocity which may not even register on accelerometer measurements. Additionally, as the overall cruising speed increases for the class of high performance aircraft, it becomes difficult to determine shallow turns since the rate of turn is inversely proportional to the forward speed of the vehicle. The higher performance aircraft cruise at high speeds and perform coordinated shallow turns, which may not register in the turn indicator algorithm, and the algorithm may cause the gyro to erect out of such shallow turns resulting in larger than expected errors.

In this embodiment, a primary processor monitors inputs to identify the existence of GPS or airdata sensor information. When GPS or airdata sensor information is available, the primary processor parses this information and uses velocity or speed data from these sensors in the attitude algorithm. In the event GPS or airdata sensor information is not available, the attitude algorithm reverts to a standard, unaided algorithm.

Referring to FIG. 13, this alternative embodiment includes the solid-state accelerometers 9, 10, 11, inertial elements 13, 14, 15, magnetic sensors 18 a, 18 b, 18 c, temperature sensor 17 coupled to an A/D converter 21 which is coupled to a processor 23 as described above with reference to FIG. 2. To provide for aiding from external sensors, the processor 23 is adapted to accept inputs from an external aiding sensor 1310, and optionally, a remote magnetometer 1300. The external aiding sensor 1310 provides airspeed or velocity such as may be obtained from an airdata measurement unit or global positioning system.

Additionally, the processor 23 may be implemented using a single processor or multiple processors. For example, two DSP processors may be used for improving processing efficiency related to the intensive Kalman filter model. When two processors are used, a primary processor calculates the attitude trajectory and Kalman filter correction estimates, and a secondary processor samples the sensor data at a very high rate, and performs digital filtering on the data. The primary processor also performs system control monitoring and external communications. The user accesses the computed data or raw sensor data digitally through a digital serial link coupled to the primary processor.

The Kalman filter, which estimates the system error parameters and gyro bias states, runs in the primary processor, for example, a floating-point processor. The aiding algorithms used by the Kalman filter to enhance performance during high dynamic maneuvers, or when used in high performance aircraft are described below.

The aiding algorithm uses a velocity or speed measurement provided by the external aiding sensor 1310 from which an inertial speed is determined. Since the speed determined from these measurements is valid along the forward direction of the vehicle, it may be used to affect the pitch measurement residual gain calculation but not the roll. Additionally, the speed measurement may be used for both the roll and pitch noise gain calculations since these two states are highly coupled.

Referring to FIG. 14, the DiffSpeedGain2 flag 1430 is based on the inertial speed measurement 1400. Inertial speed 1400 is differentiated 1410 and passed through a very low frequency cutoff high pass filter 1420 to create a smooth identifier of true dynamic acceleration changes with significant time profiles. For example, the minimum update rate of the external velocity data may be 1 Hz. The roll and pitch gyro bias portion of the state noise covariance will be scaled using the DiffSpeedGain2 flag 1420 to reduce any roll and pitch gyro bias mismodeling, explained further below. When Inertial Speed is present, the adaptive gain will be made equal to DiffSpeedGain2, but during the initialization period, the adaptive gain will be set to 1.0. If Inertial Speed is not present or if GPS and airdata stop communicating then the adaptive gain calculation will be performed as previously described herein.

FIG. 15 illustrates a shallow turn aiding algorithm using speed from, for example, a global positioning system or airdata measurement unit. The aiding algorithm is used for shallow turns, and may be disabled when the turn indicator algorithm indicates a turn is occurring. Thus, the aiding algorithm compensates for shallow turn situations in which the turn indicator algorithm is unable to determine that a turn is in progress. To prevent incorrect use during non-coordinated turn conditions such as those mainly present during ground runway operations, the algorithm determines 1500 whether speed is present. If speed is not present, the yaw rate is obtained 1522 and filtered 1541 and the algorithm determines 1532 whether the turn is coordinated. When airspeed is present, the algorithm determines 1510 whether the vehicle is airborne. If the vehicle is not airborne, the yaw rate is obtained 1520, and the algorithm determines 1530 the turn conditions by bypassing the sluggish filtering step. In this case, the aiding algorithm is no longer applied. When the vehicle is airborne, the airspeed will be greater than 40 knots. In this situation, the yaw rate is obtained 1521 and filtered 1540, and the turn conditions are determined 1531.

When speed is determined 1500 to be present, and the flight regime has been determined 1510, the airspeed and filtered yaw rate measurements are used to generate a centripetal acceleration correction to the tangential acceleration vector used in generating the attitude residuals. The algorithm is presented below. As observed in the equation, only the y-axis is affected by this centripetal correction, and hence only the roll channel is affected by this improvement.

$\begin{matrix} {{ACC}_{TAN} = {{CB}\; 2\; T*{ACC}_{BODY}}} & \left( {{Eq}.\mspace{14mu} 24} \right) \\ {{ACC}_{TAN} = \begin{bmatrix} {ACC}_{{TAN}\; X} \\ {{ACC}_{{TAN}\; Y} + {{YawRateFiltered}*{Airspeed}}} \\ {ACC}_{{TAN}\; Z} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 25} \right) \end{matrix}$

The measurement model for the Kalman filter contains components that are nonlinear in nature. The actual measurements are defined in an attitude perturbation model similar to the attitude perturbation quaternion state model described above. The transfer to attitude angle perturbations lends itself to a straightforward derivation of the angle errors by comparison to the reference accelerometer and magnetometer data available. The measurement noise covariances are defined from the performance of the accelerometers and magnetometers and are contained in R_(meas). They are implicitly made up of two separate definitions for measurement noise, one for the perturbed quaternion estimate, which directly corresponds to the accelerometer and magnetometer references, and the other for the gyro bias estimate, which can be modeled by long term observation of gyro performance. The following relationship describes the Kalman filter measurement model:

$\begin{matrix} {y_{meas} = {{C_{meas}*\delta\; x_{est}} + R_{meas}}} & \left( {{Eq}.\mspace{11mu} 26} \right) \\ {y_{meas} = {{\begin{bmatrix} {\delta\;{roll}_{ref}} \\ {\delta\;{pitch}_{ref}} \\ {\delta\;{yaw}_{ref}} \end{bmatrix}\begin{bmatrix} {\delta\;{roll}_{est}} \\ {\delta\;{pitch}_{est}} \\ {\delta\;{yaw}_{est}} \end{bmatrix}} = {\begin{bmatrix} {ACCY}_{{TAN}\;{residual}} \\ {ACCX}_{{TAN}\;{residual}} \\ {Heading}_{residual} \end{bmatrix} - \begin{bmatrix} {f_{1}\left( {\delta\; q} \right)} \\ {f_{2}\left( {\delta\; q} \right)} \\ {f_{3}\left( {\delta\; q} \right)} \end{bmatrix}}}} & \left( {{Eq}.\mspace{14mu} 27} \right) \\ {{\begin{bmatrix} {ACCY}_{{TAN}\;{residual}} \\ {ACCX}_{{TAN}\;{residual}} \\ {Heading}_{residual} \end{bmatrix} - \begin{bmatrix} {f_{1}\left( {\delta\; q} \right)} \\ {f_{2}\left( {\delta\; q} \right)} \\ {f_{3}\left( {\delta\; q} \right)} \end{bmatrix}} = {{C_{meas}*\begin{bmatrix} {\delta\;\overset{\_}{q}} \\ g_{b} \end{bmatrix}} + \begin{bmatrix} G_{\delta\;\overset{\_}{q}} \\ G_{g_{b}} \end{bmatrix}}} & \left( {{Eq}.\mspace{14mu} 28} \right) \end{matrix}$

The attitude reference error measurements are direct measurements of the Euler angle errors, and are therefore a nonlinear combination of the quaternion perturbation states. They may be obtained by mathematically rotating the measured accelerometer signals with reference to the body into the tangent or level frame, and then calculating the attitude reference error by observing any residual non-level acceleration terms in the tangent and assigning the attitude error measurements based on the magnitude of the residual terms. The accelerometer data may be filtered to remove high frequency vibration effects. The heading reference error may be obtained by calculating the heading direction as measured from the leveled magnetometers (leveling is achieved from using the CB2G matrix which is the direction cosine matrix made up of system roll and pitch only), and comparing this heading to the current estimated yaw angle obtained from the attitude trajectory. The heading error measurement then is based on the magnitude of the residual angle error difference between the magnetometer heading and yaw. Both these reference signals are derived in the following relationship:

$\begin{matrix} {{ACC}_{TAN} = {{CB}\; 2T*{ACC}_{BODY}}} & \left( {{Eq}.\mspace{14mu} 29} \right) \\ {\begin{bmatrix} {ACCX}_{{TAN}\;{residual}} \\ {ACCY}_{{TAN}\;{residual}} \\ {Heading}_{residual} \end{bmatrix} = \begin{bmatrix} {{{sign}\left( {ACC}_{{TAN}\; X} \right)}*\theta\; c_{({ADAPT})}} \\ {{- {{sign}\left( {ACC}_{{TAN}\; Y} \right)}}*\phi\; c_{({ADAPT})}} \\ {{{sign}\left( {Heading}_{ERR} \right)}*\psi\; c_{({ADAPT})}} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 30} \right) \\ {{Heading}_{ERR} = {\psi_{({yaw})} - {Heading}_{Mag}}} & \left( {{Eq}.\mspace{14mu} 31} \right) \\ {{Heading}_{Mag} = {a\;\tan\; 2\left( {{MAGY}_{TAN},{MAGX}_{TAN}} \right)}} & \left( {{Eq}.\mspace{14mu} 32} \right) \\ {\begin{bmatrix} {MAGX}_{TAN} \\ {MAGY}_{TAN} \\ {MAGZ}_{TAN} \end{bmatrix} = {\quad{{CB}\; 2\; G*\begin{bmatrix} {MAGX}_{BODY} \\ {MAGY}_{BODY} \\ {MAGZ}_{BODY} \end{bmatrix}}}} & \left( {{Eq}.\mspace{14mu} 33} \right) \end{matrix}$

The fixed angle channel corrections represent the maximum residual the Kalman filter will see upon every state update and state correction. This method assures that the Kalman filter state estimate will remain stable, and that the attitude perturbations can never grow unbounded. The channel correction derivation algorithm is presented by the relationships shown below. The magnetometer and accelerometer magnitude parameters (AccMag and MagMag) used in the noise covariance algorithm are also used in the derivation of the channel corrections, and are defined herein. The accelerometer parameter is calculated slightly differently and is shown below. During initialization period, the fixed angle channel corrections will be set to a static large value, which will provide the filter with more authority to speed up state estimate convergence. When airdata is present the ACCParam2 parameter will be calculated using the DiffAirspeed calculation defined in the above section, and employed to scale the pitch residual.

$\begin{matrix} {{{AccParam} = {\mathbb{e}}^{{- {AccMag}^{2}}*200}},{{{AccParam}\; 2} = {\mathbb{e}}^{{- {DiffAirspeed}^{2}}*2}}} & \left( {{Eq}.\mspace{14mu} 34} \right) \\ {\begin{bmatrix} {RollChannelFixedCorrection} \\ {PitchChannelFixedCorrection} \\ {YawChannelFixedCorrection} \end{bmatrix} = {\quad\begin{bmatrix} {{TMINROLL} + {\left( {{TMAXROLL} - {TMINROLL}} \right)*{AccParam}}} \\ {{TMINPITCH} + {\left( {{TMAXPITCH} - {TMINPITCH}} \right)*\begin{matrix} {AccParam}_{({NoAirdata})} \\ {AccParam}_{({WithAirdata})} \end{matrix}}} \\ {{TMINYAW} + {\left( {{TMAXYAW} - {TMINYAW}} \right)*{MagMag}}} \end{bmatrix}}} & \left( {{Eq}.\mspace{14mu} 35} \right) \\ {\left. {{if}\mspace{14mu}({CoordinatedTurn})}\Rightarrow\begin{bmatrix} {RollChannelFixedCorrection} \\ {PitchChannelFixedCorrection} \\ {YawChannelFixedCorrection} \end{bmatrix} \right. = \begin{bmatrix} {TMINTURNROLL} \\ {TMINTURNPITCH} \\ {TMINTURNYAW} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 36} \right) \\ {\left. {{if}\mspace{14mu}({KalmanFilterInitializationPhase})}\Rightarrow\begin{bmatrix} {RollChannelFixedCorrection} \\ {PitchChannelFixedCorrection} \\ {YawChannelFixedCorrection} \end{bmatrix} \right. = \begin{bmatrix} {TCALROLL} \\ {TCALPITCH} \\ {TCALYAW} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 37} \right) \end{matrix}$

The quaternion perturbation functions defined in the Kalman filter measurement model are derived from the cosine rotation matrix definition. The estimated perturbation quaternion defines a cosine rotation matrix, from which the perturbed attitude angles may be obtained and are shown below in Eq. 38-42. The elements of the cosine rotation matrix that are used to obtain the perturbed attitude angles are calculated from the corresponding estimated perturbation quaternion. Then the trigonometric definition of the attitude angles are used to define the estimated perturbed attitude angles.

$\begin{matrix} {\begin{bmatrix} {\delta\;{roll}_{est}} \\ {\delta\;{pitch}_{est}} \\ {\delta\;{yaw}_{est}} \end{bmatrix} = {\begin{bmatrix} {f_{1}\left( {\delta\; q} \right)} \\ {f_{2}\left( {\delta\; q} \right)} \\ {f_{3}\left( {\delta\; q} \right)} \end{bmatrix} = \begin{bmatrix} {a\;\tan\; 2\left( {{\tan\; 1},{\tan\; 2}} \right)} \\ {a\;{\sin\left( {2.0*\left( {{\delta\; q_{0}*\delta\; q_{2}} - {\delta\; q_{1}*\delta\; q_{3}}} \right.} \right.}} \\ {a\;\tan\; 2\left( {{\tan\; 3},{\tan\; 4}} \right)} \end{bmatrix}}} & \left( {{Eq}.\mspace{14mu} 38} \right) \\ {\mspace{79mu}{{\tan\; 1} = {2.0*\left( {{\delta\; q_{2}*\delta\; q_{3}} + {\delta\; q_{1}*\delta\; q_{0}}} \right)}}} & \left( {{Eq}.\mspace{14mu} 39} \right) \\ {\mspace{79mu}{{\tan\; 2} = {1.0 - {2.0*\left( {{\delta\; q_{2}*\delta\; q_{2}} + {\delta\; q_{1}*\delta\; q_{1}}} \right)}}}} & \left( {{Eq}.\mspace{14mu} 40} \right) \\ {\mspace{79mu}{{\tan\; 3} = {2.0*\left( {{\delta\; q_{1}*\delta\; q_{2}} + {\delta\; q_{3}*\delta\; q_{0}}} \right)}}} & \left( {{Eq}.\mspace{14mu} 41} \right) \\ {\mspace{79mu}{{\tan\; 4} = {1.0 - {2.0*\left( {{\delta\; q_{2}*\delta\; q_{2}} + {\delta\; q_{3}*\delta\; q_{3}}} \right)}}}} & \left( {{Eq}.\mspace{14mu} 42} \right) \end{matrix}$

The measurement matrix C_(meas) is calculated as:

$\begin{matrix} {C_{meas} = \begin{bmatrix} {{2*\delta\; q_{0}} - \frac{2*\delta\; q_{1}^{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{3}} - \frac{2*\delta\; q_{1}*\delta\; q_{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{2}} - \frac{2*\delta\; q_{1}*\delta\; q_{3}}{\delta\; q_{0}}} & 0_{1 \times 3} \\ {{{- 2}*\delta\; q_{3}} - \frac{2*\delta\; q_{1}*\delta\; q_{2}}{\delta\; q_{0}}} & {{2*\delta\; q_{0}} - \frac{2*\delta\; q_{2}^{2}}{\delta\; q_{0}}} & {{{- 2}*\delta\; q_{1}} - \frac{2*\delta\; q_{2}*\delta\; q_{3}}{\delta\; q_{0}}} & 0_{1 \times 3} \\ {{{- 2}*\delta\; q_{2}} - \frac{2*\delta\; q_{1}*\delta\; q_{3}}{\delta\; q_{0}}} & {{{- 2}*\delta\; q_{1}} - \frac{2*\delta\; q_{2}*\delta\; q_{3}}{\delta\; q_{0}}} & {{{- 2}*\delta\; q_{0}} - \frac{2*\delta\; q_{3}*\delta\; q_{3}}{\delta\; q_{0}}} & 0_{1 \times 3} \end{bmatrix}} & \left( {{Eq}.\mspace{14mu} 43} \right) \end{matrix}$

This matrix is the traditional Jacobian linearization used in Kalman filtering when the state estimate is defined to be a nonlinear function of the measurements. The state estimate is the perturbation quaternion, and the measurements are the reference residuals that define the observed attitude errors. Obtaining the matrix differential of each measurement linearizes the quaternion representation of the cosine rotation matrix, and is used as the first half of the measurement matrix. The second half is made up of zero elements, which shows that the gyro bias state estimate is not dependent on the actual attitude errors, but rather on the change in attitude error.

Therefore, the apparatus and processes according to the present invention provide a low-cost sensor assembly for platform stabilization systems and for other dynamic positioning and guidance control systems in automotive, marine, and aeronautical applications that require convenient gravity reference. An aiding system method is presented to provide accurate attitude determinations throughout all flight regimes.

APPENDIX A Sensor Compensation Raw Sensor Inputs ab[3] Accelerations uncorrected (ab[1] = x, ab[2] = y, ab[3] = z ωb[3] Rate Sensor uncorrected (ωb[1] = x, ωb[2] = y, ωb[3] = z) Corrected Sensor Outputs ac[3] Accelerations corrected ωc[3] Rate Sensor corrected Calibration coefficients ba[3] accelerometer bias sa[3] accel scale error L2[3] accel non-linearity bω[3] rate bias sω[3] rate scale error ma[12] misalignment table Accelerometer Channel Error al[1] = ((L2[1]*ab[1] + sa[1]*ab[1] + ba[1]) + ab[1] al[2] = ((L2[2]*ab[2] + sa[2]*ab[2] + ba[2]) + ab[2] al[3] = ((L2[3]*ab[3] + sa[3]*ab[3] + ba[3]) + ab[3] Gyro Channel Error ωl[1] = (sω[1]* ωb[1] + bω[1] + ωb[1] ωl[2] = (sω[2]* ωb[2] + bω[2] + ωb[2] ωl[3] = (sω[3]* ωb[3] + bω[3] + ωb[3] Accelerometer Compensation for Misalignment ac[1] = ma[1]*al[2] + ma[2]*al[3] + al[1]; ac[2] = ma[4]*al[1] + ma[3]*al[3]*al[2]; ac[3] = ma[5]*al[1] + ma[6]*al[3] + al[3]; Gyro compensation for misalignment ωc[1] = ma[7]* ωl[2] + ma[8]* ωl[3] + ωl[1] ωc[2] = ma[10]* ωl[1] + ma[9]* ω[3] + ωl[2] ωc[3] = ma[11]* ωl[I] + ma[12]* ωl[2] + ω1[3]

APPENDIX B Factory Calibration alev[3] = level frame acceleration/tilt of platform ac[3] = compensated body frame acceleration readings see Step 2 dc[3][3] = direction cosines matrix alev[1] = dc[1][1] * ac[1] + dc[1][2] * ac[2] + dc[1][3]*ac[3]; alev[2] = dc[2][1] * ac[1] + dc[2][2] * ac[2] + dc[2][3]*ac[3]; alev[3] = dc[3][1] * ac[1] + dc[3][2] * ac[2] + dc[3][3]*ac[3];

APPENDIX C Update Quaternion and Normalize Quaternion DT = Time change in seconds from last update divided by 2 DQ = Normalization coefficient a4, b4, c4, d4 = temporary quaternion a, b, c, d = quaternion representation of attitude ωc[3] = angular rate sampled over DT interval by A/D converter      (1, 2, 3 = X, Y, Z respectively) ωcx = corrective rate signals x generated in Appendix A, para. 7 ωcy = corrective rate signals y generated in Appendix A, para. 7 ωcz = corrective rate signal z (azimuth) /*compute temporary quaternion as a function of sensed rates and   previous quaternion */ a4 = DT* ((ωc[3] + ωcz)*b − (ωc[2] + ωcy)*c + (−1*ωc[1] + ωcx)*d); b4 = DT* ((−1*ωc[3] − ωcz)*a + ωc[1] + ωcx)*c + (ωcy − ωc[2]*d); c4 = DT* ((ωc[2] + ωcy)*a − (ωc[1] + ωcx)*b + (−1*ωc[3] + ωcz)*d); d4 = DT* ((ωc[1] − ωcx)*a + (ωc[2] − ωcy)*b + (ωc[3] − ωcz)*c); /* update quaternion */ a += a4; b += b4; c += c4; d += d4; /* normalize quaternion */ DQ = 1 − 05*(a*a + b*b + c*c + d*d − 1); a *= DQ; b *= DQ; c *= DQ; d *= DQ;

APPENDIX D Convert Quaternion to Direction Cosines Matrix d1, d2, d3, c11, c12, c13, c14, c22, c23, c24, c33, c34 Temporary storage dc[3][3] 3 × 3 direction cosines matrix /* compute temporary storage */ d1 = a + a; d2 = b + b; d3 = c + c; c11 = d1 * a; c12 = d1 * b; c13 = d1 * c; c14 = d1 * d; c22 = d2 * b; c23 = d2 * c; c24 = d2 * d; c33 = d3 * c; c34 = d3 * d; /* update direction cosines */ dc[1][1] = 1 − c22 − c33; dc[2][2] = 1 − c11 − c33; dc[3][3] = 1 − c11 − c22; dc[2][1] = c12 − c34; dc[1][3] = c13 − c24; dc[3][2] = c23 − c14; dc[1][2] = c12 + c34; dc[3][1] = c13 + c24; dc[2][3] = c23 + c14;

APPENDIX E Generate Corrective Rates Option 1: Proportional Gain ωcx = −KG * alev[2]; ωcy = KG * alev[1]; Option 2: Non-linear Gain if (alev[2] > 0.0) ωcx = −1*UG else ωcx = UG if(alex[1] > 0.0) ωcy = UG; else ωcy = −1*UG

APPENDIX F Heading/Azimuth Corrective Rate ωcz: azimuth corrective rates ct: cosine of true heading st: sine of true heading ωcz = KG * (ct*dc[2][1] − st*dc[1][1])

APPENDIX G Extract Euler Angle for Direction Cosines Roll, Pitch, Yaw—final outputs in Euler Angle format Roll = atan (dc[3][2]/dc[3][3]) Pitch = asin (dc[3][1]) Heading = atan (dc[3][2], dc[1][1]) 

1. A method for correcting a predicted attitude of an accelerating object, the method comprising: receiving external aiding data; calculating an inertial speed from the external aiding data; adjusting a sensor correction factor in response to the inertial speed; and, correcting the predicted attitude of the accelerating object in response to the adjusted sensor correction factor.
 2. The method of correcting the predicted attitude of claim 1, wherein receiving external aiding data comprises: receiving a calculated velocity measurement.
 3. The method of correcting the predicted attitude of claim 1, wherein receiving external aiding data comprises: receiving an airspeed measurement.
 4. The method of correcting the predicted attitude of claim 1, wherein adjusting the sensor correction factor in response to the inertial speed comprises scaling a pitch measurement residual gain in response to the inertial speed.
 5. The method of correcting the predicted attitude of claim 1, wherein adjusting the sensor correction factor in response to the inertial speed comprises scaling a roll bias in response to the inertial speed.
 6. The method of correcting the predicted attitude of claim 1, wherein adjusting the sensor correction factor in response to the inertial speed comprises scaling a pitch bias in response to the inertial speed.
 7. A system for correcting a predicted attitude of an accelerating object, comprising: a processor for receiving external aiding data and computing an inertial velocity; and, an adaptive filter, coupled to the processor, comprising a sensor correction factor adjusted in response to the inertial velocity, for predicting the attitude of the accelerating object.
 8. A system for correcting the predicted attitude of claim 7, wherein the external aiding data is a velocity measurement.
 9. A system for correcting the predicted attitude of claim 7, wherein the external aiding data is an airspeed measurement.
 10. A system for correcting the predicted attitude of claim 7, wherein the adaptive filter is a Kalman filter.
 11. A system for correcting the predicted attitude of claim 7, wherein the sensor correction factor is a pitch measurement residual gain.
 12. A system for correcting the predicted attitude of claim 7, wherein the sensor correction factor is a roll bias.
 13. A system for correcting the predicted attitude of claim 7, wherein the sensor correction factor is a pitch bias. 